EP2697399B1 - Alloy, magnet core and process for producing a strip made of an alloy - Google Patents

Description

The present invention relates to an alloy, in particular a soft magnetic alloy suitable for use as a magnetic core, a magnetic core and a method for producing an alloy strip. Nanocrystalline alloys based on a composition Fe _100-abcdxyz Cu _a Nb _b M _c T _d Si _x B _y Z _z can be used as a magnetic core in various applications. The US 7,583,173 discloses a wound magnetic core used inter alia in a current transformer consisting of (Fe _1-a Ni _a ) _100-xyzabc Cu _x Si _y B _z Nb _α M ' _β M'' _γ where a ≤0.3 , 0.6 ≤ x ≤ 1.5, 10 ≤ y ≤ 17, 5 ≤ z ≤ 14, 2 ≤ α ≤ 6, β ≤ 7, γ ≤ 8, M 'at least one of V, Cr, Al and Zn and M "is at least one of C, Ge, P, Ga, Sb, In, and Be.

The EP 0 271 657 A2 also discloses alloys with a summary on this basis.

The EP 1 045 402 discloses an amorphous alloy in the form of a strip 25 mm wide and 18 μm thick. The tape is heat treated under tension and has a grain size of less than 50 nm, the remanence ratio is less than 10%.

These alloys, also in the form of tapes, can be used as a magnetic core in various components, such as power transformers, current transformers, and storage chokes.

For magnetic core applications, the lowest possible production costs are generally desirable. However, the cost reduction should have as little or no effect on the operation of the magnetic core.

In some applications of magnetic cores, further reduction of the size and weight of the magnetic core is desirable so that the size and weight of the component itself can be further reduced. At the same time, however, no increase in the manufacturing cost of the magnetic core is desired.

The object is therefore to provide an alloy which is suitable for use as a magnetic core, which can be produced more cheaply. Another object is to select the alloys so that the size and / or weight of the magnetic core can be reduced compared to a conventional magnetic core.

This is solved by the subject matters of the independent claims. Further developments are the subject of the respective dependent claims.

_{According to the} invention, an alloy is specified which consists of Fe _100-abcdxyz Cu _a Nb _b M _c T _d Si _x B _y Z _z and up to 1 atom% of impurities. M is one or more of Mo, Ta or Zr, T is one or more of V, Mn, Cr, Co or Ni, Z is one or more of C, P or Ge and 0 at% ≤ a <1.5 Atom%, 0 atom% ≦ b <2 atom%, 0 atom% ≦ (b + c) <2 atom%, 0 atom% ≦ d <5 atom%, 10 atom% <x <18 atom%, 5 atom% <y <11 at% and 0 at% <z <2 at%. The alloy is further formed in the form of a band and has a nanocrystalline structure in which at least 50% by volume of the grains have an average size of less than 100 nm. The alloy also has a hysteresis loop with a central linear part, a remanence ratio, J _{r /} J _s , <0.1, and a ratio of coercive force, H _c , to anisotropic field strength, H _a , <10%.

The alloy thus has a composition with a niobium content of less than 2 atomic percent. This has the advantage that the raw material costs are lower compared to a composition with a higher niobium content, since niobium is a relatively expensive element. Further, the lower limit of the silicon content and the upper limit of the boron content of the alloy are determined so that the alloy can be made in the form of a strip under tension in a continuous furnace, thereby achieving the above-mentioned magnetic properties. Consequently, with this manufacturing method, the alloy, despite the lower niobium content, can also have the desired soft magnetic properties for magnetic core applications.

The shape as a band not only makes it possible to manufacture the alloy under tension in a continuous furnace, but also to manufacture a magnetic core having any number of windings. Consequently, the size and magnetic properties of the magnetic core can be easily adjusted by appropriate selection of the windings to the application. Due to the nanocrystalline structure with a particle size of less than 100 nm in at least 50% by volume of the alloy, a low saturation magnetostriction is achieved at high saturation polarization. The heat treatment under tensile stress, with suitable alloy selection, results in a magnetic hysteresis loop with a central linear part, a remanence ratio of less than 0.1 and a coercive field strength of less than 10% of the anisotropy field. Linked to this are low re-magnetization losses and permeability, which is independent of the applied magnetic field or bias in the linear, central part of the hysteresis loop, which are desired in magnetic cores for applications such as current transformers, power transmitters and storage chokes.

Herein, the central part of the hysteresis loop is defined as the part of the hysteresis loop that lies between the anisotropy field strength points that characterize the transition to saturation. A linear part of this central part of the hysteresis loop is defined herein by a nonlinearity factor NL of less than 3%, the nonlinearity factor being calculated as follows: $$\mathit{NL}\left(\mathrm{in}\%\right)=100\left(\delta J_{\mathrm{on}}+\delta J_{\mathrm{from}}\right)/\left(2J_{\mathrm{s}}\right)$$

In this case, δJ _on or δJ _{ab designate} the standard deviation of the magnetization from a compensation straight line by the ascending or descending branch of the hysteresis loop between magnetization values of ± 75% of the saturation polarization J _s .

This alloy is thus particularly suitable for a magnetic core, which has a reduced size and a smaller weight at lower raw material costs and at the same time the desired soft magnetic properties for use as a magnetic core.

In one embodiment, the remanence ratio of the alloy is less than 0.05. The hysteresis loop of the alloy is thus even more linear or flatter. In another embodiment, the ratio of coercive force to anisotropic field strength is less than 5%. Also is In this embodiment, the hysteresis loop even more linear, so that the Ummagnetisierungsverluste are even lower.

In one embodiment, the alloy further has a permeability μ of 40 to 3000 or 80 to 1500. In another embodiment, the alloy has a permeability between about 200 and 9000. In these and other examples, the permeability is determined primarily by the choice of tensile stress in the heat treatment. The tensile stress can be up to about 800 MPa without the band breaking. Thus, with a given composition, it is possible to cover a band having a permeability within the entire permeability range from μ = 40 to about μ = 10000. Especially linear loops result in the range of low permeabilities, i. in about μ = 40 to 3000.

Such relatively low permeabilities are advantageous for current transformers, power transmitters, storage chokes, and other applications in which the magnetic core should not become ferromagnetically saturated so that the inductance does not suffer when high electrical currents flow through windings around the magnetic core.

Suitable permeability ranges result from the specific requirements of the respective application. Suitable ranges are 1500 to 3000, 200 to 1500 and 50 to 200. For example, for DC-DC current transformers, a permeability μ of about 1500 to about 3000 is advantageous, while for power transmitters a permeability range of about 200 to 1500 and for storage chokes rather a permeability range of about 50 to 200 is particularly suitable.

The lower the permeability, the higher the electrical currents through the windings of the magnetic core can be without saturating the material. Likewise, with the same permeability, these currents can be higher, the higher the saturation polarization, J _s , of the material. On the other hand, the inductance of the magnetic core increases with the permeability and the size. In order to build magnetic cores with simultaneously high inductance and high current tolerance, it is therefore advantageous to use alloys with higher saturation polarization. For example, in one embodiment, by reducing the niobium content, the saturation polarization of J _s = 1.21 T is increased to J _s = 1.34 T, ie, more than 10%. This can ultimately be exploited without sacrificing the size and weight of the core to reduce.

The alloy may have a saturation magnetostriction of less than 5 ppm in magnitude. Alloys with a saturation magnetostriction below these limits have particularly good soft magnetic properties even with internal stress, especially when the permeability is not significantly greater than 500. For higher permeabilities it is advantageous to select alloys with smaller values of saturation magnetostriction.

The alloy may also have a saturation magnetostriction of less than 2 ppm, preferably less than 1 ppm. Alloys with a saturation magnetostriction below these limits have particularly good soft magnetic properties even with internal stress, in particular if the permeability μ is greater than 500 or greater than 1000. In one embodiment, the alloy is niobium-free, ie, b = 0. This embodiment has the advantage that the raw material costs are even further reduced since the element niobium is completely omitted.

In another embodiment, the alloy is copper-free, i. a = 0. In another embodiment, the alloy is niobium and copper free, i. a = 0 and b = 0.

In further embodiments, the alloy comprises niobium and / or copper, where 0 <a ≦ 0.5 and 0 <b ≦ 0.5.

In further embodiments, the silicon content and / or the boron content is further defined such that the alloy has 14 atom% <x <17 atom% and / or 5.5 atom% <y <8 atom%.

As already mentioned above, the alloy has the shape of a band. This band may have a thickness of 10 microns to 50 microns. This thickness makes it possible to wind a magnetic core with a large number of windings, which at the same time has a small outer diameter.

In a further embodiment, at least 70% by volume of the grains have an average size of less than 50 nm. This allows a further increase in the magnetic properties.

The alloy is heat-treated in the form of a ribbon under tension to produce the desired magnetic properties. The alloy, ie the finished heat-treated strip, is thus also characterized by a structure which originated by this manufacturing process. In one embodiment, the crystallites have an average size of about 20-25 nm and a remanent elongation in the tape longitudinal direction between about 0.02% and 0.5%, which is proportional to the tensile stress applied during the heat treatment. For example, a heat treatment under a tensile stress of 100 MPa results in an elongation of about 0.1%.

The crystalline grains may have an elongation of at least 0.02% in a preferred direction.

An alloy magnetic core according to any one of the above embodiments is also given. The magnetic core may be in the form of a wound tape, wherein to form the magnetic core, depending on the application, the tape may be wound in a plane or as a solenoid about an axis.

The band of the magnetic core may be coated with an insulating layer to electrically insulate the windings of the magnetic core from each other. The layer may be, for example, a polymer layer or a ceramic layer. The tape may be coated with the insulating layer before and / or after winding into a magnetic core.

As already mentioned, the magnetic core according to one of the preceding embodiments can be used in various components. There is also provided a power transformer, a current transformer, and a storage reactor having a magnetic core according to one of these embodiments.

A method for producing a tape is also _{disclosed which comprises} : an amorphous alloy tape having a composition consisting of Fe _100-abcdxyz Cu _a Nb _b M _c T _d Si _x B _y Z _z and up to 1 Atom% impurities, where M is one or more of the elements Mo, Ta or Zr, T one or more of the elements V, Mn, Cr, Co or Ni and Z one or more of the elements C, P or Ge and 0 atom% ≤ a <1.5 atom%, 0 atom% ≦ b <2 atom%, 0 atom% ≦ (b + c) <2 atom%, 0 atom% ≦ d <5 atom%, 10 atom% <x <18 atom %, 5 atom% <y <11 atom% and 0 atom% ≦ z <2 atom%. This tape is heat-treated under tension in a continuous furnace at a temperature T _a , where 450 ° C ≤ Ta ≤ 750 ° C.

This composition can be prepared with a heat treatment between 450 ° C and 750 ° C under tension with suitable magnetic properties for use as a magnetic core. The heat treatment results in the formation of a nanocrystalline microstructure in which at least 50% by volume of the grains have an average size smaller than 100 nm. In particular, this composition having less than 2 atomic percent of niobium can be prepared by this method to have a hysteresis loop with a central linear part, a remanence ratio, J _{r /} J _s , <0.1, and a coercive force ratio, H _c , to anisotropic field strength, H _a , <10%.

The strip is heat treated in the pass. Consequently, the belt is pulled through the continuous furnace at a speed s. This speed s can be adjusted so that a residence time of the strip in a temperature zone of the continuous furnace with the temperature within 5% of the temperature T _a is between 2 seconds and 2 minutes. In this case, the time to heat the tape to the temperature T _{a is of a} comparable order of magnitude as the duration of the heat treatment itself. The same applies to the duration of the subsequent cooling. This residence time leads in this tempering temperature range to the desired structure and the desired magnetic properties.

In one embodiment, the tape is pulled through the continuous furnace under a tension of between 5 and 160 MPa. In another embodiment, the tape is pulled through the continuous furnace under a tensile stress of 20 MPa to 500 MPa. It is also possible to pull the tape through the oven with a higher tension up to about 800 MPa without tearing it. This range of tensile stress is suitable for achieving the desired magnetic properties in the above-mentioned compositions.

The value of the permeability μ achieved is inversely proportional to the tensile stress σ _a applied during the heat treatment. In order to achieve a predetermined value of the relative permeability μ, a tensile stress σ _{a is} required during the heat treatment which satisfies the relationship σ _a ≈ α / μ. In one embodiment, α has a value of α ≈ 48,000 MPa. In another embodiment, α has a value of, for example, α ≈ 36,000 MPa. Thus, values in the range α ≈ 30000 MPa to α ≈ 70000 MPa can be used for the alloys according to the invention and the corresponding heat treatment process. The exact value of α depends on the composition, the tempering temperature and to some extent on the tempering time.

ausgewählt.The tensile stress that leads to the desired magnetic properties may therefore be dependent on the composition of the alloy and on the tempering temperature as well as the tempering time. In one exemplary embodiment, the tensile stress σ _a required for a given permeability μ is determined from the permeability μ _{test of} a _test annealing under a tensile stress σ _test according to the relationship $${\mathrm{\sigma }}_{\mathrm{a}}\approx {\mathrm{\sigma }}_{\mathrm{TEST}}{\mu }_{\mathrm{TEST}}/\mu$$

selected.

The desired magnetic properties may also be dependent on the tempering temperature T _a and consequently set by the selection of the tempering temperature. In one embodiment, the temperature T _{a is selected} depending on the niobium content b according to the relationship (T _x1 + 50 ° C) ≦ T _a ≦ (T _x2 + 30 ° C). In this case, T _x1 and T _x2 correspond to the crystallization temperatures defined by the maximum of the heat of transformation, which are determined by means of thermal standard methods such as DSC (differential scanning calometry) at a heating rate of 10 K / min.

In a further embodiment, a desired value of the permeability or anisotropic field strength, as well as a permitted deviation range is predetermined. In order to achieve this value over the length of the belt, magnetic properties of the belt are continuously measured when leaving the continuous furnace. When deviations are detected from the allowed deviation ranges of the magnetic properties, the tension on the belt is adjusted accordingly to bring the measured values of the magnetic properties back within the allowable deviation ranges. This embodiment reduces the deviations of the magnetic properties over the length of the tape, so that the magnetic properties within a magnetic core are more homogeneous and / or the magnetic properties of a plurality of magnetic cores made of a single tape deviate less. Thus, the uniformity of the soft magnetic properties of the magnetic cores, especially in commercial production, can be improved.

Figur 1

zeigt ein Diagramm von Hystereseschleifen von Vergleichsbeispielen nanokristallinem Fe_77-xCu₁Nb_xSi_15.5B_6.5 mit unterschiedlichem Niobgehalt nach Wärmebehandlung in einem Magnetfeld quer zur Bandrichtung,

Figur 2

zeigt ein Diagramm von Hystereseschleifen von nanokristallinem Fe_77-xCu₁Nb_xSi_15.5B_6.5 nach Wärmebehandlung unter einer Zugspannung längs der Bandrichtung für unterschiedliche Niobgehalte,

Figur 3

zeigt ein Diagramm des Remanenzverhältnisses von nanokristallinem Fe_77-xCu₁Nb_xSi_15.5B_6.5 nach Wärmebehandlung im Magnetfeld und nach Wärmebehandlung unter Zugspannung als Funktion des Nb-Gehaltes,

Figur 4

zeigt ein Diagramm der Sättigungspolarisation von Fe_77-xCu₁Nb_xSi_15.5B_6.5 als Funktion des Nb-Gehaltes,

Figur 5

zeigt ein Diagramm von Sättigungsmagnetostriktion λ _s, Anisotropiefeld H _a, Koerzitivfeldstärke H _c, Remanenzverhältnis J _r/J _s und Nichtlinearitätsfaktor NL von Fe_75.5Cu₁Nb_1.5Si_15.5B_6.5 nach Wärmebehandlung unter einer Zugspannung bei unterschiedlichen Anlasstemperaturen,

Figur 6

zeigt ein Diagramm von Remanenzverhältnis J _t/J _s und Koerzitivfeldstärke H _c der Legierung Fe₇₇Cu₁Si_15.5B_6.5 nach Wärmebehandlung unter einer Zugspannung,

Figur 7

zeigt das mittels Differential Scanning Calometry mit einer Aufheizrate von 10 K/min gemessene Kristallisationsverhalten der Legierung Fe₇₇Cu₁Si_15.5B_6.5 und die Definition der Kristallisationstemperaturen T _x1 und T _x2,

Figur 8

zeigt die Röntgenbeugungsdiagramme für die Legierung Fe₇₇Cu₁Si_15.5B_6.5 im amorphen Ausgangszustand und nach Wärmebehandlung unter Zug bei verschiedenen Anlasstemperaturen entsprechend unterschiedlichen Kristallisationsstufen.

Figur 9

zeigt ein Diagramm von Permeabilität µ, Anisotropiefeld H _a, Koerzitivfeldstärke H _c, Remanenzverhältnis J _r/J _s und Nichtlinearitätsfaktor NL von nanokristallinem Fe_75.5Cu₁Nb_1.5Si_15.5B_6.5 nach Wärmebehandlung unter der angegebenen Zugspannung σ _a,

Figur 10

zeigt die untere und obere optimale Anlasstemperatur T _a1 und T _a2 für verschiedene Legierungszusammensetzungen als Funktion Kristallisationstemperaturen T _x1 und T _x2.

Figur 11

zeigt ein Diagramm von Koerzitivfeldstärke H _c und Remanenzverhältnis J _r/J _s der Legierung Fe₈₀Si₁₁B₉ und eine Vergleichszusammensetzung Fe_78.5Si₁₀B_11.5 nach einer Wärmebehandlung unter einer Zugspannung,

Figur 12

zeigt ein Diagramm von Hystereseschleifen einer Legierung Fe₈₀Si₁₁B₉ und eine Vergleichszusammensetzung Fe_78.5Si₁₀B_11.5 nach Wärmebehandlung unter unterschiedlichen Zugspannungen, und

Figur 13

zeigt eine schematische Ansicht eines Durchlaufofens.

Tabelle 1

zeigt den Nichtlinearitätsfaktor NL für verschiedene Nb-Gehalte der Legierung Fe_77-xCu₁Nb_xSi_15.5B_6.5 nach Wärmebehandlung im Magnetfeld (Vergleichsbeispiel)und nach Wärmebehandlung unter einer mechanischen Zugspannung (erfindungsgemäßes Verfahren),

Tabelle 2

zeigt gemessene Kristallisationstemperaturen und geeignete Anlasstemperaturen T _a für Anlasszeiten von etwa 2s bis 10s für verschiedene Nb-Gehalte der Legierung Fe_77-xCu₁Nb_xSi_15.5B_6.5,

Tabelle 3

zeigt magnetische Eigenschaften einer Legierung Fe₇₆Cu₁Nb_1.5Si_13.5B₈ nach Wärmebehandlung im Durchlauf bei 610°C unter einer Zugspannung von ca. 120 MPa als Funktion der Anlasszeit t _a,

Tabelle 4

zeigt magnetische Eigenschaften einer Legierung Fe₇₆Cu_0.5Nb_1.5Si_15.5B_6.5 nach Wärmebehandlung mit der angegebenen Zugspannung σ _a,

Tabelle 5

zeigt im Herstellzustand gemessene Sättigungspolarisation J _s, nach Wärmebehandlung bei unterschiedlichen Anlasstemperaturen T _a gemessene Werte von Nichtlinearität NL, Remanenzverhältnis J _r/J _s, Koerzitivfeldstärke H _c, Anisotropiefeldstärke H _a und relative Permeabilität µ verschiedener Legierungszusammensetzungen,

Tabelle 6

zeigt im Herstellzustand gemessene Sättigungspolarisation J _s, nach Wärmebehandlung gemessene Werte von Nichtlinearität NL, Remanenzverhältnis J _r/J _s, Koerzitivfeldstärke H _c, Anisotropiefeldstärke H _a und relative Permeabilität µ verschiedener Legierungszusammensetzungen, und

Tabelle 7

zeigt die Sättigungsmagnetostriktion λ _s verschiedener Legierungszusammensetzungen gemessen im Herstellzustand und nach Wärmebehandlung unter Zug bei der angegebenen Anlasstemperatur T _a.

Embodiments will now be explained in more detail with reference to the following examples, tables and drawings.

FIG. 1

shows a diagram of hysteresis loops of comparative examples of nanocrystalline Fe _77-x Cu ₁ Nb _x Si _15.5 B _6.5 with different niobium content after heat treatment in a magnetic field transverse to the ribbon direction,

FIG. 2

shows a diagram of hysteresis loops of nanocrystalline Fe _77-x Cu ₁ Nb _x Si _15.5 B _6.5 after heat treatment under a tensile stress along the ribbon direction for different niobium contents,

FIG. 3

shows a graph of the remanence ratio of nanocrystalline Fe _77-x Cu ₁ Nb _x Si _15.5 B _6.5 after heat treatment in the magnetic field and after heat treatment under tensile stress as a function of the Nb content,

FIG. 4

shows a diagram of the saturation polarization of Fe _77-x Cu ₁ Nb _x Si _15.5 B _6.5 as a function of the Nb content,

FIG. 5

shows a plot of saturation magnetostriction λ _s , anisotropy field H _a , coercive force H _c , remanence ratio J _r / J _s and nonlinearity factor NL of Fe _75.5 Cu ₁ Nb _1.5 Si _15.5 B _6.5 after heat treatment under tensile stress at different tempering temperatures,

FIG. 6

shows a diagram of remanence ratio J _t / J _s and coercive force H _{c of} the alloy Fe ₇₇ Cu ₁ Si _15.5 B _6.5 after heat treatment under a tensile stress,

FIG. 7

shows the crystallization behavior of the alloy Fe ₇₇ Cu ₁ Si _15.5 B _6.5 measured by differential scanning calometry at a heating rate of 10 K / min and the definition of the crystallization _temperatures T _x1 and T _x2 ,

FIG. 8

shows the X-ray diffraction diagrams for the alloy Fe ₇₇ Cu ₁ Si _15.5 B _6.5 in the amorphous initial state and after heat treatment under tension at different tempering temperatures corresponding to different crystallization stages.

FIG. 9

shows a diagram of permeability μ , anisotropy field H _a , coercive force H _c , remanence ratio J _r / J _s and nonlinearity factor NL of nanocrystalline Fe _75.5 Cu ₁ Nb _1.5 Si _15.5 B _6.5 after heat treatment under the specified tensile stress σ _a ,

FIG. 10

shows the lower and upper optimum tempering temperatures T _a1 and T _a2 for various alloy compositions as a function of crystallization _temperatures T _x1 and T _x2 .

FIG. 11

shows a diagram of coercive force H _c and remanence ratio J _r / J _{s of} the alloy Fe ₈₀ Si ₁₁ B ₉ and a comparative _composition Fe _78.5 Si ₁₀ B _11.5 after a heat treatment under a tensile stress,

FIG. 12

shows a diagram of hysteresis _{loops of} an alloy Fe ₈₀ Si ₁₁ B ₉ and a comparative _composition Fe _78.5 Si ₁₀ B _11.5 after heat treatment under different tensile stresses, and

FIG. 13

shows a schematic view of a continuous furnace.

Table 1

shows the nonlinearity factor NL for various Nb contents of the alloy Fe _77-x Cu ₁ Nb _x Si _15.5 B _6.5 after heat treatment in the magnetic field (comparative example) and after heat treatment under a mechanical tensile stress (method according to the invention),

Table 2

shows measured crystallization temperatures and suitable tempering temperatures T _a for tempering times of about 2s to 10s for different Nb contents of the alloy Fe _77-x Cu ₁ Nb _x Si _15.5 B _6.5 ,

Table 3

shows magnetic properties of an alloy Fe ₇₆ Cu ₁ Nb _1.5 Si _13.5 B ₈ after heat treatment in the pass at 610 ° C under a tensile stress of about 120 MPa as a function of the tempering time t _a ,

Table 4

shows magnetic properties of an alloy Fe ₇₆ Cu _0.5 Nb _1.5 Si _15.5 B _6.5 after heat treatment with the specified tensile stress σ _a ,

Table 5

shows saturation polarization J _s measured in the production state, values of non-linearity NL, remanence ratio J _r / J _s , coercive field strength H _c , anisotropic field strength H _a and relative permeability μ of different alloy compositions measured after heat treatment at different tempering temperatures T _a .

Table 6

shows saturation polarization J _s measured in the manufacturing state, values of non-linearity NL, remanence ratio J _r / J _s , coercive force H _c , anisotropic field strength H _a and relative permeability μ of various alloy compositions measured after heat treatment

Table 7

shows the saturation magnetostriction λ _{s of} various alloy compositions measured in the state of manufacture and after heat treatment under tension at the specified tempering temperature T _a .

FIG. 1 shows a diagram of hysteresis loops of nanocrystalline alloys in the form of a band.

The investigations were carried out by way of example on 6 mm and 10 mm wide and typically 17 μm to 25 μm thick metal strips. However, the inventive idea is not limited to these dimensions.

The bands have a composition of Fe _77-x Cu ₁ Nb _x Si _15.5 B _6.5 . The hysteresis loops are measured after heat treatment in the magnetic field, wherein a heat treatment of 0.5 h at 540 ° C in a magnetic field of H = 200 kA / m is performed transversely to the belt direction. FIG. 1 shows that with decreasing Nb content the hysteresis loops become non-linear. This nonlinear hysteresis loop is undesirable in some magnetic core applications because the core loss losses are increased.

Table 1 shows the nonlinearity factors NL of the hysteresis loops shown in Figs. 1 and 2 for various heat treatments and various Nb contents. In particular, Table 1 shows the nonlinearity factor of nanocrystalline Fe _77-x Cu ₁ Nb _x Si _15.5 B _6.5 after heat treatment in the magnetic field for 0.5 h at a temperature of 540 ° C and after a heat treatment under tensile stress of 100 MPa for 4 s at 600 ° C for different Nb contents.

FIG. 3 shows a graph of the remanence ratio J _r / J _s heat-treated samples as a function of Nb content. In particular shows FIG. 3 the remanence ratio of nanocrystalline Fe _77-x Cu ₁ Nb _x Si _15.5 B _6.5 after heat treatment in the magnetic field of 0.5 h at temperatures of 480 ° C to 540 ° C and after a heat treatment under tensile stress of 4 s at temperatures between 520 ° C and 700 ° C as a function of Nb content.

For a heat treatment in the magnetic field, with open circular symbols in the FIG. 3 is shown, especially linear loops with a remanence ratio smaller than 0.1 and a nonlinearity factor smaller than 3% are reliably achieved only for Nb contents greater than 2 at%. In contrast to For example, for a heat treatment under tensile stress, linear loops having a remanence ratio less than 0.1 and a non-linearity factor less than 3% can be reliably achieved for Nb contents less than 2 at% and even for compositions without niobium.

From the results of FIGS. 1 and 3 It can be seen that a minimum Nb content of preferably greater than 2 at% is required to produce a tape having suitable magnetic properties for magnetic core application when the heat treatment is performed in a magnetic field.

Tables 1 to 6 and the FIGS. 2 to 12 show that low remanence ratio linear loops can be achieved with compositions having a niobium content of less than 2 atomic% when the heat treatment is under a belt lengthwise mechanical tension. These compositions have the advantage that raw material costs are reduced since niobium is a relatively expensive element.

FIG. 2 shows a diagram of hysteresis loops of bands after heat treatment in the run with an effective tempering time of 4s at a temperature of 600 ° C and under a tensile stress of about 100 MPa.

As starting time in the run, the time is defined at which the band passes through the temperature zone at which the temperature within 5% corresponds to the tempering temperature given here. In this case, the time to heat the tape to the tempering temperature is comparable to the duration of the heat treatment itself. The same applies to the duration of the subsequent cooling.

FIG. 2 shows that for Nb contents less than 2 at%, hysteresis loops with a central linear part and a small remanence ratio can be obtained. The composition with Nb 3at% is a comparative example and the compositions with Nb <2at% are examples according to the invention. The arrow shows by way of example the definition of the anisotropy field strength H _a .

FIG. 3 FIG. 3 is a graph of a remanent ratio comparison for such tension tempered samples as shown in FIG FIG. 3 are shown with filled diamonds, and for magnetic field annealed samples shown with open circle symbols as a function of Nb content. Alloys with Nb contents below 2 at% have a small remanence ratio of less than 0.05 only when heat-treated under tension. However, when these compositions are annealed under a magnetic field, the remanence ratio is significantly higher, so that these alloys are not suitable for some magnetic core applications. Even for the alloy Fe ₇₇ Cu ₁ Si _15.5 B _6.5, ie without addition of Nb, a substantially linear loop with a remanence ratio of less than 0.05 results when heat-treated under a tensile stress.

FIG. 4 shows a plot of the saturation polarization of alloys with a composition of Fe _77-x Cu ₁ Nb _x Si _15.5 B _6.5 as a function of the Nb content. The alloys with reduced Nb content have a significantly increased saturation polarization. This can be beneficial in a corresponding weight and Reduced manufacturing costs of the magnetic core can be implemented. Thus, in addition to reduced raw material costs, a further advantage results since the device having the magnetic core can be made smaller.

FIG. 5 shows a diagram of saturation magnetostriction λ _s , anisotropy field H _a , coercive force H _c , remanence ratio J _r / J _s and nonlinearity factor NL of a composition Fe _75.5 Cu ₁ Nb _1.5 Si _15.5 B _6.5 after heat treatment of about 4 seconds duration under a tensile stress of approx. 50 MPa as a function of the tempering temperature. The anisotropy field H _a corresponds to the field in which the linear part of the hysteresis loop passes into saturation, which in the FIG. 2 is shown.

The tempering temperatures, between which the desired properties can be achieved, are in the range of about 535 ° C to 670 ° C, which is highlighted hatched in the figure.

The hatched area shows the area in which linear loops with small saturation magnetostriction, high anisotropy field and small remanence ratio result. This is also the area in which the alloys have particularly linear loops. In the embodiment of FIG. 5 Thus, the most suitable tempering temperature between 535 ° C and 670 ° C.

These temperature limits are largely independent of the magnitude of the tensile stress. However, they depend on the duration of the heat treatment and the Nb content. For example, they decrease with decreasing Nb content or with prolonged heat treatment off, as in the FIG. 6 and Table 2.

FIG. 6 shows the starting behavior of a niobium-free alloy variant, in which the optimal tempering temperatures in the range of about 500 ° C to 570 ° C, ie significantly lower than the composition of FIG. 5 lie. In particular shows FIG. 6 a diagram of the remanence ratio J _t / J _s and the coercive force H _{c of} the alloy Fe ₇₇ Cu ₁ Si _15.5 B _6.5 after heat treatment for 4 seconds at T _a = 613 ° C under a tensile stress of about 50 MPa. The optimum tempering temperatures according to the invention here are in the range of about 500 ° C to 570 ° C. This yields, as indicated schematically by the inset, a flat linear hysteresis loop with a remanence ratio of less than 0.1.

FIG. 7 shows the crystallization behavior measured by differential scanning calometry (DSC) at a heating rate of 10 K / min using the example of the alloy Fe ₇₇ Cu ₁ Si _15.5 B _6.5 . One recognizes two crystallization stages which are characterized by the crystallization _temperatures T _x1 and T _x2 . The temperature range limited by T _{x 1} and T _x2 in the DSC measurement corresponds to the range of optimum tempering temperatures which corresponds to this FIG. 6 for the alloy is between 500 ° C and 570 ° C.

FIG. 8 shows the X-ray diffraction diagrams for the alloy Fe ₇₇ Cu ₁ Si _15.5 B _6.5 in the amorphous initial state and after heat treatment under tension at different tempering temperatures corresponding to the different crystallization _stages defined by T _x1 and T _x2 . In particular shows FIG. 8 the X-ray diffraction pattern after a heat treatment under tension for 4s at 515 ° C, ie in the starting area, where magnetic properties according to the invention are achieved, and at 680 ° C, ie in the unfavorable starting area where no linear hysteresis loops with a small remanence ratio can be achieved more.

From the analysis of the diffraction maxima, it follows that at tempering temperatures where linear hysteresis loops with a small remanence ratio result, essentially only cubic Fe-Si crystallites form, which are embedded in an amorphous minority matrix, as the crystalline phase. In the case of the alloy Fe ₇₇ Cu ₁ Si _15.5 B _6.5 , the average size of these crystallites is approximately in the range 38-44 nm. If an analogous analysis is carried out with the alloy composition Fe _75.5 Cu ₁ Nb _1.5 Si _15.5 B _6.5 corresponding optimal tempering temperatures an average crystallite size in the range 20-25 nm.

In the second stage of crystallization, boride phases crystallize out of the residual amorphous matrix, which adversely affect the magnetic properties and lead to a non-linear loop with a high remanence ratio and high coercive force.

Table 2 shows further examples, as well as supplementary data in the form of the differential scanning calorimetry (DSC) at 10K / min measured crystallization _temperatures T _x1 , which corresponds to the crystallization of bcc-FeSi, and T _x2 , which corresponds to the crystallization of borides , The suitable tempering temperature is approximately between T _x1 and T _x2 and leads to a structure of nanocrystalline grains with a mean grain size less than 50 nm, which in an amorphous Embedded matrix, and the desired magnetic properties.

However, T _x1 and T _x2 and the tempering temperatures T _a depend on the heating rate and the duration of the heat treatment. Therefore, with a heat treatment time of less than 10 seconds, the optimum tempering temperatures at higher temperatures than the differential scanning calorimetry (DSC) at 10K / min measured crystallization temperatures T _x1 and T _x2 of Table 2. Accordingly, for longer tempering times, for example, 10 min up to 60 minutes, the optimum tempering temperatures T _a typically 50 ° C to 100 ° C lower than the values of T _a listed in Table 2 for a heat treatment time of a few seconds.

Accordingly, the tempering temperatures T _a depending on the composition and duration of the heat treatment according to the doctrine of FIG. 5 and optionally adjusted according to the crystallization temperatures measured in the DSC according to Table 2.

Table 3 shows the influence of tempering time on the example of the alloy composition Fe ₇₆ Cu ₁ Nb _1.5 Si _13.5 B ₈ . For tempering times in the range of a few seconds to a few minutes hardly a significant influence on the resulting magnetic properties is shown. This applies as long as the tempering temperature T _{a is} between the limit temperatures discussed with reference to Table 2. The latter amount in the present embodiment T _x1 = 489 ° C and T _x2 = 630 ° C from the DSC measurement at 10 K / min or T _a1 = 540 ° C and T _a2 = 640 ° C for a heat treatment of 4 s duration ,

The tempering temperature in the present embodiment is T _a = 610 ° C and thus lies between the lower and upper values of both definitions of limit temperatures. The crystallization temperatures measured at a heating rate of 10 K / min correspond approximately to the optimum starting range for an isothermal heat treatment of a few minutes duration.

FIG. 9 shows the dependence of the permeability, the anisotropy field, the coercive field strength, the remanence ratio and the nonlinearity factor on the tensile stress applied during the heat treatment. In particular, FIG. 9 shows a diagram of the permeability, the anisotropy field, the coercive field strength, the remanence ratio and the nonlinearity factor of nanocrystalline
Fe _75.5 Cu ₁ Nb _1.5 Si _15.5 B _6.5 after heat treatment for 4 seconds at 613 ° C under the specified tensile stress σ _a . In all cases, this resulted in a remanence ratio of typically less than J _r / J _s <0.04 and a nonlinearity factor of less than 2%.

Table 4 shows another example of the dependence of permeability, anisotropy field, coercive force, remanence ratio and non-linearity factor on the tensile stress applied during the heat treatment. In particular, the table shows the permeability, anisotropy field, coercivity, remanence ratio and nonlinearity factor of nanocrystalline Fe ₇₆ Cu _0.5 Nb _1.5 Si _15.5 B _6.5 after heat treatment for 4 seconds at 605 ° C under the given tensile stress σ _a . In all cases, this resulted in a remanence ratio of typically less than J _r / J _s <0.1 and a nonlinearity factor of less than 3%.

FIG. 9 and Table 4 show that the anisotropic field strength H _a and the permeability μ can be adjusted in _a targeted manner by adjusting the tensile stress σ _a . In order to achieve a predetermined value of the anisotropic field strength H _a or permeability μ , a tensile stress σ _a ≈ α μ ₀ H _a / J _s or σ _a ≈ α / μ is required during the heat treatment, where μ ₀ = (4π 10 ^-7 Vs / (Am)) denotes the magnetic field constant. Here, α denotes a material parameter which may depend primarily on the alloy composition, but also on the tempering temperature and tempering time. Typical values are in the range of α ≈ 30,000 MPa to α ≈ 70,000 MPa. In particular, results for the example in FIG. 9 a value of α ≈ 48000 MPa and for the example in Table 3 a value of α ≈ 36000 MPa.

The embodiments in FIG. 9 and Table 3 also show that the smaller the set permeability, the more linear the loops can be achieved. Thus, for permeabilities less than about μ = 3000, particularly linear loops with a nonlinearity of less than 2% and a remanence ratio J _r / J _s <0.05 result.

Cu

0≤ a < 1.5,

Nb

0 ≤ b < 2,

• M eines oder mehrere der Elemente Mo, Ta, oder Zr mit 0 ≤ b+c
• < 2 ist,
• T eines oder mehrere der Elemente V, Mn, Cr, Co oder Ni mit 0 ≤ d < 5 ist,

Si

10 < x < 18

B

5 < y < 11

Z eines oder mehrere der Elemente C, P oder Ge mit 0 ≤ z < 2,
wobei die Legierung bis zu 1 Atom% Verunreinigungen aufweisen kann. Typische Verunreinigungen sind C, P, S, Ti, Mn, Cr, Mo, Ni, und Ta.The bands of the preceding embodiments comprise an alloy having the composition
Fe _100-abcdxyz Cu _a Nb _b M _c T _d Si _x B _y Z _z where

Cu

0≤a <1.5,

Nb

0 ≤ b <2,

• M one or more of the elements Mo, Ta, or Zr with 0 ≤ b + c
• <2 is,
• T is one or more of the elements V, Mn, Cr, Co or Ni with 0 ≦ d <5,

Si

10 <x <18

B

5 <y <11

Z is one or more of the elements C, P or Ge with 0 ≦ z <2,
wherein the alloy may have up to 1 atom% impurities. Typical impurities are C, P, S, Ti, Mn, Cr, Mo, Ni, and Ta.

The composition can exert an influence on the magnetic properties in certain heat treatments. In order to achieve the desired magnetic properties in a composition, the heat treatment and in particular the tensile stress can be adjusted.

Table 5 shows examples of the alloy, which were approximately 4 seconds heat-treated under a tension of 50 MPa at an optimum for the respective composition tempering temperature T _A, and a Comparative Example having a composition with a niobium content of above 2 atomic%. The remaining examples, numbered 1 to 10, represent compositions according to the invention having an Nb content of less than 2 at%. FIG. 10 shows in addition the optimum tempering temperatures and the crystallization temperatures of the alloy examples 1 to 10. In particular shows FIG. 10 the lower and upper optimum tempering temperatures T _a1 and T _a2 for a tempering time of 4 s as a function of the crystallization temperatures T _x1 and T _x2 measured in the DSC at 10 K / min.

• Fe_71.5Co_2.5Ni_0.5Cr_0.5V_0.5Mn_0.2Cu_0.7Nb_0.5Mo_0.5Ta_0.4Si_15.5B_6.5C_0.2

in 20 µm Banddicke und 10 mm Bandbreite hergestellt. Die Legierung weist eine Sättigungspolarisation von J _s = 1.25 T auf und reagiert auf Wärmebehandlung unter Zugspannung ähnlich wie z.B. die Legierungsbeispielen 2 - 5 aus Tabelle 3. So ergibt sich bei einer etwa 4 s dauernden Wärmebehandlung bei 600°C unter einer Zugspannung von 50 MPa ein Nichtlinearitätsfaktor von 0.4%, ein Remanenzverhältnis J _r/J _s = 0.01, eine Koerzitivfeldstärke von H _c = 6 A/m, ein Anisotropiefeld von H _a = 855 A/m und ein Permeabilitätswert von µ = 1160.These examples show that for alloys according to the invention the composition can be varied within certain limits. Within the previously indicated limits (1) instead of Nb further elements such as Mo, Ta and / or Zr (2) instead of iron other transition metals such as V, Mn, Cr, Co and or Ni or (3) elements such as C, P and / or Ge can be added without the properties change significantly. To substantiate this, as another embodiment, the alloy composition

• Fe _71.5 Co _2.5 Ni _0.5 Cr _0.5 V _0.5 Mn _0.2 Cu _0.7 Nb _0.5 Mo _0.5 Ta _0.4 Si _15.5 B _6.5 C _0.2

manufactured in 20 μm strip thickness and 10 mm strip width. The alloy has a saturation polarization of J _s = 1.25 T and reacts to heat treatment under tensile stress similar to, for example, the alloy examples 2-5 in Table 3. Thus results in a heat treatment of about 4 s at 600 ° C under a tensile stress of 50 MPa a non-linearity factor of 0.4%, a remanence ratio J _r / J _s = 0.01, a coercive field strength of H _c = 6 A / m, an anisotropy field of H _a = 855 A / m and a permeability value of μ = 1160.

From Table 5 shows that even without addition of Cu desirable magnetic properties.

Table 6 therefore shows other examples of alloys in which the Cu content was varied systematically and a heat treatment of about 7 seconds duration was carried out at 600 ° C under a tensile stress of about 15 MPa. Specifically, in Table 6, the element Fe was gradually replaced by Cu, with the remaining alloying components remaining unchanged.

Table 6 shows no significant influence of the Cu content on the magnetic properties for Cu contents below 1.5at%. However, the addition of Cu promotes the Embrittlement tendency of the strips during production. In particular, alloys with Cu contents greater than 1.5at% (such as the alloy no. 15 from Table 6) already in the production state a strong embrittlement, so that a 20 .mu.m thick band of alloy Fe _74.5 Cu ₂ Nb _1.5 Si _15.5 B _6.5 at a bending diameter of about 1 mm can break.

Such a brittle belt can not be caught or wound up directly during the casting process due to the high production line speeds (25-30 m / s) after leaving the cooling roller or only with great difficulty during the casting process. This makes the tape production uneconomical. Also, such break even at the beginning of brittle bands in the heat treatment to an increased extent, especially before they enter the zone of elevated temperature. With such a break, the heat treatment process is interrupted and the tape must be threaded through the oven again.

On the other hand, alloys with a Cu content of less than 1.5at% can be bent to a bending diameter of twice the strip thickness, ie typically less than 0.06 mm, without breaking. This allows the tape to be rewound directly during casting. Furthermore, the heat treatment of such initially ductile bands is much easier. Alloys with a Cu content of less than 1.5 at% become embrittled only after the heat treatment, but only after they have left the furnace and are cooled again. The probability of a ligament tear during the heat treatment is thus significantly lower. Also, in most cases, belt transport through the oven can continue despite demolition. All in all, ductile tapes can thus be produced more easily and thus more economically, as well as heat-treated at first.

The compositions shown in Tables 5 and 6 are nominal at% compositions which, within an accuracy of typically ± 0.5 at%, are consistent with the individual element concentrations found in the chemical analysis.

The silicon content and the boron content also exert an influence on the magnetic properties of this type of nanocrystalline alloy with a niobium content of less than 2 atomic% when made under tensile stress.

The examples from Tables 3 to 6 have the following desired combination of properties, ie a linear magnetization loop in the central part with a remanence ratio J _r / J _s <0.1 and a small coercive force H _c which is typically only a few percent of the anisotropic field strength H _a ,

The Figures 11 and 12 compare the magnetic properties of the compositions Fe ₈₀ Si ₁₁ B ₉ and Fe _78.5 Si ₁₀ B _11.5 . FIG. 11 shows a plot of the course of coercive force H _c and remanence ratio J _r / J _{s of} both alloys after heat treatment under a tensile stress of about 50 MPa as a function of the tempering temperature T _a . The coercive field strength H _c and the remanence ratio J _r / J _{s of} the alloy Fe ₈₀ Si ₁₁ B ₉ according to the invention is represented by filled circle symbols and the comparative _composition Fe _78.5 Si ₁₀ B _{11.5 shown} by open triangular symbols, after a heat treatment of 4 seconds duration at the tempering temperature T _a under a tensile stress of about 50 MPa.

FIG. 12 shows a diagram of hysteresis loops of the two alloys after heat treatment for 4s at about 565 ° C under tensile stresses of 50 MPa (dashed line) and 220 MPa (solid line). The hysteresis loop of the alloy Fe ₈₀ Si ₁₁ B _{9 according to} the invention is shown on the left and that of the comparative _composition Fe _78.5 Si ₁₀ B _11.5 is shown on the right.

Although in the Figures 11 and 12 The alloys shown differ only slightly in their chemical composition, resulting in such large differences in the magnetic properties of both alloys.

Thus, the composition of the invention Fe ₈₀ Si ₁₁ B ₉ after heat treatment between about 530 ° C and 570 ° C, a linear magnetization loop with a small remanence ratio J _r / J _s <0.1 and a low coercive force, which is well below 100 A / m and ultimately only a few percent of the anisotropic field strength H _a .

_{By contrast} , the composition Fe _78.5 Si ₁₀ B _{11.5 has} a high remanence ratio throughout the entire heat treatment range. Even the lowest values of the remanence ratio, which are achieved at tempering temperatures between 540 ° C and 570 ° C, are still around J _r / J _s ≈ 0.5 (see. Fig. 11 ). Furthermore, at these lowest values of J _r / J _s, an unfavorably high coercive field strength of approximately H _c ≈ 800-1000 A / m results. As a result, loses the central part of the magnetization loop to linearity and the strong split of the hysteresis loop leads to disadvantageous high Ummagnetisierungsverlusten (see. Fig. 12 ).

These embodiments show that for alloy compositions having a Si content of greater than 10 at% and a B content of less than 11 at% after heat treatment under tensile stress, a flat, substantially linear hysteresis loop with a remanence ratio J _r / J _s < 0.1 and a low coercive field strength, which is well below 100 A / m and not more than 10% of the anisotropy field. With a lower silicon content and a higher boron content than these limits, the desired magnetic properties are not achieved in this tensile stress treatment.

The upper limit of the Si content and the lower limit of the boron content are also examined. While the alloy composition Fe ₇₅ Cu _0.5 Nb _1.5 Si _17.5 B _5.5 (see Alloy No. 5 of Table 5) could be easily prepared as an amorphous ductile tape and had desirable properties after heat treatment, the alloy composition had Fe ₇₅ Cu _0.5 Nb _1.5 Si ₁₈ B ₅ after heat treatment only borderline magnetic properties and the alloy composition Fe ₇₅ Cu _0.5 Nb _1.5 Si _18.5 B _4.5 could no longer be produced as a ductile amorphous band.

These embodiments show that for alloy compositions having a Si content of less than 18 at% and a B content of more than 5 at% after heat treatment under tensile stress, a flat, substantially linear hysteresis loop with a remanence ratio J _r / J _s < 0.1 and a low coercive field strength, which is well below 100 A / m and not more than 10% of the anisotropy field. At a silicon content higher than 18 at% and a boron content lower than 5at%, the desired magnetic properties in this tensile heat treatment are not reaches or can no longer produce an amorphous and ductile band.

Table 7 shows the saturation magnetostriction constant λ _{s of} various alloy compositions measured in the state of manufacture and after a heat treatment of 4 _seconds under a tension of 50 MPa at the indicated tempering temperature T _a . In particular, an annealing temperature was selected which is not more than 50 ° C. away from the maximum possible tempering temperature T _a2 , since in this way particularly small values of the magnetostriction are obtained for a given composition (cf. FIG. 5 ), which are ultimately determined by the alloy composition. The effect of the Si content of the alloy is shown.

Table 7 shows in addition to FIG. 5 in that, after heat treatment under tensile stress, a significant reduction of the saturation magnetostriction results, which can lead to reproducible magnetic properties. In particular, little or no influence of mechanical stresses on the hysteresis loop results with small magnetostriction. Such mechanical stresses can occur when the heat-treated tape is wound into a magnetic core, or when the magnetic core is embedded in a trough or plastic mass or subsequently provided with wire turns for further protection. From this it is possible to derive particularly advantageous compositions, namely those with a small magnetostriction.

As evidenced by the examples of Table 7, particularly advantageous magnetostriction values of less than 5 ppm can be achieved if the Si content is greater than 13 at% and the heat treatment temperature is not more than 50 ° C is below the upper limit T _{a2 of} the optimal starting range. Even smaller values of the saturation magnetostriction, which are smaller than 2 ppm in absolute value, can be achieved if the Si content is greater than 14 at% and less than 18 at%, and the heat treatment temperature is not more than 50 ° C. below the upper limit T _{a2 of} the optimum tempering range lies. Even smaller values of the saturation magnetostriction, which are smaller than 1 ppm in absolute terms, can be achieved if the Si content is greater than 15 at% and and the heat treatment temperature is not more than 50 ° C. below the upper limit T _{a2 of} the optimum tempering range.

A small amount of magnetostriction is the more important the higher the permeability. Thus, alloys with a permeability greater than 500, or greater than 1000 have a comparatively low dependence on mechanical stresses when the saturation magnetostriction is less than 2 ppm or less than 1 ppm in absolute terms.

The alloy may also have a saturation magnetostriction of less than 5 ppm in magnitude. Alloys with a saturation magnetostriction below these limits still have good soft magnetic properties even at internal stress, when the permeability is less than 500.

The value of the saturation magnetostriction may still slightly depend on the tensile stress σ _a applied during the heat treatment. For example, for alloy Fe _75.5 Cu ₁ Nb _1.5 Si _15.5 B _6.5 at a heat treatment of 4s at 610 ° C the following values are obtained: λ _s ≈ 1 ppm at σ _a ≈ 50 MPa, λ _s ≈ 0.7 ppm σ _a ≈ 260 MPa and λ _s ≈ 0.3 ppm at σ _a ≈ 500 MPa This corresponds to a small decrease the magnetostriction of Δλ _s ≈ -0.15 ppm / 100 MPa. The other alloy compositions show similar behavior.

FIG. 13 shows a schematic view of a device 1, which is suitable to produce the alloy with a composition according to one of the preceding embodiments in the form of a band. The apparatus 1 comprises a continuous furnace 2 with a temperature zone 3, this temperature zone being set so that the temperature in the furnace in this zone is within 5 ° C. of the tempering temperature T _a . The device 1 further comprises a coil 4, on which the amorphous alloy 5 is wound, and a take-up spool 6, on which the heat-treated belt 7 is received. The tape is drawn at a speed s from the spool 4, through the continuous oven 2 to the take-up spool 6. In this case, the belt 7 is in the direction of the device 9 to the device 10 under a tensile stress σ _a .

The apparatus 1 further comprises an apparatus 8 for continuously measuring the magnetic properties of the belt 6 after it has been heat treated and drawn out of the continuous furnace 2. In the area of this device 8, the belt 7 is no longer under tension. The measured magnetic properties can be used to set the tensile stress σa under which the belt 7 is pulled through the continuous furnace 2. This is with the arrows 9 and 10 in the FIG. 13 shown schematically. By measuring the magnetic properties and continuously adjusting the tensile stress, the uniformity of the magnetic properties over the length of the tape can be improved.

Claims (15)

1. Alloy, consisting of

   Fe_{100-a-b-c-d-x-y-z}C_uaNb_bM_cT_dSi_xB_yZ_z and up to 1at% impurities, M being one or more of the elements Mo, Ta or Zr, T being one or more of the elements V, Mn, Cr, Co or Ni, Z being one or more of the elements C, P or Ge, 0at% ≤ a < 1.5at%, 0at% ≤ b < 2at%, 0at% ≤ (b+c) < 2at%, 0at% ≤ d < 5at%, 10at% < x < 18at%, 5at% < y < 11at% and 0at% ≤ z < 2at%,

   is configured in tape form,

   comprising a nanocrystalline structure in which at least 50%vol of the grains have an average size of less than 100 nm,

   a hysteresis loop with a central linear part,

   a remanence ratio Jr/Js < 0.1 and

   a ratio of coercive field strength H_c to anisotropic field strength H_a of < 10%,

   wherein the tape is producible by heat treatment under tensile stress in a continuous furnace at a temperature T_a , wherein 450°C ≤ Ta ≤ 750°C, and pulling through the continuous furnace at a speed s such that the period of time which the tape spends in a temperature zone of the continuous furnace with a temperatur T _a is between 2 seconds and 2 minutes.
2. Alloy according to claim 1, wherein the remanence ratio Jr/Js is < 0.05 and/or the ratio of coercive field strength to anisotropic field strength is < 5% and/or the alloy further comprises a permeability µ of between 40 and 3000 and/or further comprises a saturation magnetostriction of less than 2 ppm, preferably less than 1 ppm and/or the alloy comprises a permeability of less than 500 and a saturation magnetostriction of less than 5 ppm.
3. Alloy according to claim 1 or claim 2, wherein b < 0.5 and/or a < 0.5 and/or 14at% < x < 17at% and 5.5at% < y < 8at% and/or the tape commprises a thickness of 10 µm to 50 µm.
4. Alloy according to one of claims 1 to 3, wherein at least 70% of the grains comprise an average size of less than 50 nm and/or the crystalline grains comprise an elongation of at least 0.02% in a preferred direction.
5. Magnetic core made of an alloy according to one of claims 1 to 4.
6. Magnetic core according to claim 5, having the form of a wound tape.
7. Magnetic core according to claim 5 or 6, wherein the tape is coated with an insulating layer.
8. DC-tolerant current transformer comprising a magnetic core according to one of claims 5 to 7 comprising a permeability of between 1500 and 3000.
9. Power transformer comprising a magnetic core according to one of claims 5 to 7, comprising a permeability of between 200 and 1500.
10. Storage choke comprising a magnetic core according to one of claims 5 to 7, comprising a permeability of between 50 and 200.
11. Process for producing a tape comprising the following:

    providing a tape made of an amorphous alloy with a composition consisting of Fe_{100-a-b-c-d-x-y-z}Cu_aNb_bM_cT_dSi_xB_yZ_z and up to 1at% impurities, M being one or more of the elements Mo, Ta and Zr, T being one or more of the elements V, Mn, Cr, Co or Ni, Z being one or more of the elements C, P or Ge, 0at% being ≤ a < 1.5at%, 0at% ≤ b < 2 Atom%, 0at% ≤ (b+c) < 2at%, 0at% ≤ d < 5at%, 10at% < x < 18at%, 5at% < y < 11at% and 0at% ≤ z < 2at%,

    heat treating the tape under tensile stress in a continuous furnace at a temperature T_a , wherein 450°C ≤ Ta ≤ 750°C,

    wherein the tape is pulled through the continuous furnace at a speed s such that the period of time which the tape spends in a temperature zone of the continuous furnace with the temperatur T_a is between 2 seconds and 2 minutes.
12. Process according to claim 11, wherein the tape is pulled through the continuous furnace under a tensile stress of 5 MPa 800 MPa.
13. Process according to claim 11 or claim 12, the tensile stress σ_a is selected dependent on composition according to the ratio σ_a ≈ σ_Testµ_Test/µ, µ being the desired permeability and µ_Test being the permeability achieved at a test stress σ_Test.
14. Process according to one of claims 11 to 13, wherein the temperature T_a is selected dependent on the niobium content b according to the ratio (T_x1 + 50°C) ≤ Ta ≤ (Tx₂ + 30°C).
15. Process according to one of claims 11 to 24, wherein

    a desired permeability or anisotropic field value, a maximum remanence ratio Jr/Js value of less than 0.1, a maximum values of the ratio of coercive field strength to anisotropic field strength H _c /H_a of less than 10% and a permitted deviation range for each of these values is predetermined,

    magnetic properties of the tape are continuously measured as it leaves the continuous furnace, and

    if deviations from the permitted magnetic properties deviation are observed, the tensile stress at the tape is adjusted accordingly to bring the measured magnetic property values back within the permitted deviation range.

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